Tunable Mixed-Mode Voltage Differencing Buffered Amplifier-Based Universal Filter with Independently High-Q Factor Controllability

Abstract

This paper proposes the design of a mixed-mode universal biquad configuration, which realizes generic filter functions in all four possible modes, namely voltage mode (VM), current mode (CM), transadmittance mode (TAM), and transimpedance mode (TIM). The filter architecture employs two voltage differencing buffered amplifiers (VDBAs), two resistors and two capacitors, and can provide lowpass (LP), bandpass (BP), highpass (HP), bandstop (BS), and allpass (AP) biquadratic filtering responses without any circuit alteration. All passive elements used are grounded, except VM. The circuit not only allows for the electronic tuning of the natural angular frequency (ω_o), but also achieves orthogonal tunability of the quality factor (Q). It also provides the feature of availability of output voltage at the low-output impedance terminal in VM and TIM, and does not require inverting-type or double-type input signals to realize all the responses. Moreover, in all modes of operation, the high-Q filter can be easily obtained by adjusting a single resistance value. Influences of the VDBA nonidealities and parasitic elements are also discussed in detail. PSPICE simulations with TSMC 0.18-µm CMOS process parameters and experimental testing results with commercially available IC LT1228s have been used to validate the theoretical predictions.

1. Introduction

The design and synthesis of active frequency-selective filters have a very significant role in the areas of continuous-time signal processing, instrumentation and measurement applications, and wireless communication. In recent years, the design of general mixed-mode universal biquadratic filters with input voltages and/or currents and output voltages and/or currents has received a lot of attention from researchers. Considering the nature of input and output signals, the filters can be classified into four possible modes, i.e., voltage mode (VM), current mode (CM), transadmittance mode (TAM), and transimpedance mode (TIM). The VM and CM operations perform frequency filtering behavior on voltage and current signals, respectively. The TAM and TIM operations can be used as bridges for connecting a VM filter to any of the CM circuits and vice versa. Accordingly, the mixed-mode universal filters that provide all generic filtering responses in all four modes increase the versatility and flexibility of practical filtering applications and requirements. Consequently, these filters are worthy of investigation and research. Therefore, in the recent past, several structures realizing mixed-mode universal biquadratic filters with a variety of high-performance active elements have appeared in the literature [1,2,3,4,5,6,7,8,9,10,11,12,13,14,15,16,17,18,19,20,21,22,23,24,25,26,27,28,29,30,31,32,33,34,35,36,37,38,39,40,41,42,43,44,45,46].

Table 1. A comparison chart of previously related mixed-mode universal biquad filters.

Related Works/ Year	Configuration	Number of Components Used		Filter Functions Realized				Grounded Passive Elements	Inbuilt Tunability	Independent Control of ωo and Q	Need for Inverting or Double Input Signal(s)
		Active	Passive	VM	CM	TAM	TIM
[1]/2003	MISO	OTA = 6	C = 2	all five	all five	--	--	yes	yes	no	no
[2]/2003	MIMO	DO-CCCII = 4	C = 2	LP, BP, HP	LP, BP, HP	LP, BP, HP, BS	LP, BP, HP	yes	yes	yes	no
[3]/2004	MISO	CCII = 5	R = 7, C = 2	all five	all five	all five	all five	no	no	yes	no
[4]/2004	MISO	CCII = 6, DO-CCII = 1	R = 8, C = 2	all five	all five	all five	all five	no	no	yes	yes
[5]/2005	SIMO	CFOA = 4	R = 9, C = 2, switch = 1	all five	all five	all five	all five	no	no	no	no
[6]/2006	SIMO	FTFN = 3	R = 3, C = 2	LP, BP, HP	LP, BP, HP	BP, HP	LP, BP	no	no	no	no
[7]/2006	MISO	CCII = 3	R = 4, C = 2, switch = 2	all five	all five	all five	all five	no	no	no	no
[8]/2009	SIMO/MISO	FDCCII = 1	R = 3, C = 2	all five	all five	BP, HP	all five	no	no	yes	no
[9]/2009	SIMO	MO-CCCII = 5	C = 2	LP, BP, HP	LP, BP, HP	LP, BP, HP	LP, BP, HP	yes	yes	yes	no
[10]/2009	SIMO	DVCC = 3	R = 3, C = 2, MOS = 6	LP, BP, BS	all five	all five	LP, BP	yes	no	yes	no
[11]/2009	MISO	OTA = 5	C = 2	all five	all five	all five	all five	yes	yes	yes	yes
[12]/2009	MISO	MO-CCII = 3	R = 3, C = 2	--	all five	--	all five	no	no	no	no
[13]/2010	MISO	OTA = 3, DO-OTA = 1, MO-OTA = 1	C = 2	all five	all five	all five	all five	yes	yes	no	yes
[14]/2010	MISO/MIMO	DO-CCCII = 2	R = 2, C = 2	all five	all five	all five	all five	no	yes	yes	no
[15]/2010	SIMO	CCCCTA = 2	C = 2	LP, BP	all five	all five	LP, BP	no	yes	no	no
[16]/2010	MISO/MIMO	SCFOA = 1	R = 3, C = 2	all five	LP, BP, BS	--	--	no	no	no	yes
[17]/2011	SIMO	CCCCTA = 3	C = 2	LP, BP, HP	all five	all five	LP, BP, HP	yes	yes	no	no
[18]/2011	SIMO	DDCC = 3	R = 4, C = 2	all five	all five	all five	all five	no	no	yes	no
[19]/2011	MISO	MO-CCCCTA = 1	C = 2	--	all five	--	all five	yes	yes	no	no
[20]/2013	MIMO	MO-CCCII = 4	C = 2	all five	all five	all five	all five	yes	yes	no	yes
[21]/2013	MISO/MIMO	VDTA = 2	C = 2	all five	--	all five	--	no	yes	yes	no
[22]/2016	MIMO	FDCCII = 1, DDCC = 1	R = 6, C = 2	all five	all five	all five	all five	no	no	yes	yes
[23]/2016	MIMO	FDCCII = 2	R = 5, C = 2	all five	all five	all five	all five	no	no	no	no
[24]/2016	MISO/MIMO	MCCTA = 1	R = 2, C = 2	all five	all five	all five	all five	no	yes	yes	no
[25]/2016	MISO	DP-CCII = 6, MO-CCII = 2	R = 4, C = 2	all five	all five	all five	all five	yes	no	yes	yes
[26]/2016	SIMO	VDTA = 1	R = 1, C = 3	LP, BP, HP	LP, BP, HP	--	--	no	yes	yes	no
[27]/2016	SISO	DPCF = 5, VF = 2	R = 4, C = 2, switch = 3	all five	all five	all five	all five	no	yes	yes	no
[28]/2017	SIMO	CCCCTA = 3	C = 2	all five	all five	all five	LP, BP, HP	yes	yes	yes	no
[29]/2017	SIMO	VDTA = 3	C = 2	LP, BP, HP	--	all five	--	yes	yes	yes	no
[30]/2017	SIMO	OTA = 3, MO-OTA = 3	C = 2	all five	all five	all five	all five	yes	yes	no	no
[31]/2017	SIMO	DVCC = 1, MO-CCII = 1	R = 4, C = 2	--	all five	--	all five	no	no	yes	no
[32]/2017	SIMO	OTA = 1, MO-OTA = 3	C = 2, switch = 1	--	LP, BP, HP	LP, BP, HP	--	yes	yes	yes	no
[33]/2017	MISO	DXCCDITA = 1	R = 2, C = 2	all five	all five	BP, HP	all five	no	yes	no	yes
[34]/2017	MISO	DO-CCCII = 2	R = 1, C = 2	all five	all five	BP, HP	all five	no	yes	no	yes
[35]/2018	SIMO	FDCCII = 2	R = 4, C = 2	all five	all five	all five	all five	no	no	yes	no
[36]/2018	MISO	DVCC = 5	R = 5, C = 2	all five	all five	all five	all five	yes	no	yes	no
[37]/2018	SIMO	VDGA = 2	C = 3	LP, BP, HP	LP, BP, HP	--	--	no	yes	no	no
[38]/2019	SIMO	VCII = 3, I-CB = 1	R = 3, C = 3	LP, BP, HP	HP, BS, AP	LP, BP, HP	LP, BP, HP	no	no	no	no
[39]/2019	MISO	VD-DXCC = 1	R = 2, C = 2	all five	all five	--	--	no	yes	yes	yes
[40]/2020	MISO	OTA = 5	C = 2	all five	all five	all five	all five	yes	yes	yes	no
[41]/2020	MISO/MIMO	DDCC = 3	R = 4, C = 2	all five	all five	all five	all five	no	no	no	no
[42]/2020	SIMO/MISO	EXCCTA = 2	R = 4, C = 2, switch = 1	all five	all five	all five	all five	no	yes	yes	no
[43]/2020	SIMO	VDGA = 1	R = 2, C = 2	LP, BP, HP	LP, BP, HP	--	--	no	yes	yes	no
[44]/2020	MISO	VD-DDCC = 2	R = 3, C = 2	all five	--	all five	--	yes	yes	yes	no
[45]/2021	MISO/MIMO	VD-EXCCII = 1	R = 3, C = 2	all five	all five	all five	all five	no	yes	yes	no
[46]/2021	MISO/MIMO	EX-CCCII = 1	R = 1, C = 2	all five	all five	all five	BP, HP	no	yes	yes	yes
Proposed circuit	MISO/ SIMO	VDBA = 2	R = 2, C = 2	all five	all five	all five	LP, BP	yes (except for VM)	yes	yes	no

Notes: “ -- ”: not provided, MISO: multiple-input single-output configuration, MIMO: multiple-input multiple-output configuration, SIMO: single-input multiple-output configuration, SISO: single-input single-output configuration, OTA: operational transconductance amplifier, DO-OTA: dual-output OTA, MO-OTA: multiple-output OTA, DO-CCCII: dual-output second-generation current-controlled conveyor, MO-CCCII: multiple-outputs current-controlled conveyor, CCII: second-generation current conveyor, DO-CCII: dual-output CCII, MO-CCII: multiple-output CCII, FDCCII: fully differential current conveyor, CFOA: current feedback operational amplifier, SCFOA: specific CFOA, FTFN: four-terminal floating nullor, DVCC: differential voltage current conveyor, DDCC: differential difference current conveyor, VD-DDCC: voltage differencing DDCC, CCCCTA: current-controlled current conveyor transconductance amplifier, VDTA: voltage differencing transconductance amplifier, MCCTA: modified current conveyor transconductance amplifier, DXCCDITA: dual X current conveyor differential input transconductance amplifier, DP-CCII: digitally programmable current conveyor, DPCF: digitally programmable current follower, VF: voltage follower, VDGA: voltage differencing gain amplifier, VD-DXCC: voltage differencing dual X current conveyor, VCII: second-generation voltage conveyor, I-CB: inverting current buffer, EXCCTA: extra X current conveyor transconductance amplifier, VD-EXCCII: voltage differencing extra X CCII, EX-CCCII: extra X CCCII.

presents a comparative study of earlier-reported mixed-mode universal filters based on various types of high-performance active components. A deep investigation of the available literature reveals that several exemplary filter topologies introduced in [1,12,16,19,21,26,29,31,32,37,39,43,44] do not provide the different filtering responses in all four modes of operation. In [1,2,3,4,5,6,7,9,10,11,12,13,17,18,20,25,27,28,29,30,32,36,38,40,41], they require more than two active components for the design. The use of more active components results in higher power dissipation and a large chip area. Additionally, a multitude of the previously discussed mixed-mode filters [3,4,5,6,7,8,10,12,16,18,22,23,25,27,31,35,36,38,41,42,44,45] employ an excessive number (at least five) of passive components. It has been observed that the realizations of [3,4,5,6,7,8,12,14,15,16,18,21,22,23,24,26,27,31,33,34,35,37,38,39,41,42,43,45,46] still used some floating passive components, which is unfavorable from integrated circuit (IC) implementation viewpoint. To obtain various filtering responses or to change the operating mode, the designs in [5,7,27,32,42] need structural modification with a programmable switching technique. This technique needs to employ some external switches, which practically lead to increasing switching noise. The filter structures given in [3,4,5,6,7,8,10,12,16,18,22,23,25,31,35,36,38,41] do not provide the feature of inbuilt tunability of filter parameters. Furthermore, the important filter parameters, i.e., natural angular frequency (ω_o) and quality factor (Q), for the circuits [1,5,6,7,12,13,15,16,17,19,20,23,30,33,34,37,38,41] are interactive. Although the circuits of [4,13,22,25,27,30,31,32,38] allow the realization of different functions of the universal filter with the same topology, they employ two different types of active components, which are not modular, and increase the complexity of the resulting circuit. In other works [8,16,19,24,26,33,39,43,45,46], some mixed-mode universal filters based on a single active element were previously reported. However, the active devices used for these realizations are complex active components, resulting in a complicated internal structure [8,24,33,39,43,45,46]. Furthermore, the single active element-based filter circuits [16,26,39,43] function only in dual modes of operation. Therefore, it should be concluded that the filter structures presented in [1,2,3,4,5,6,7,8,9,10,11,12,13,14,15,16,17,18,19,20,21,22,23,24,25,26,27,28,29,30,31,32,33,34,35,36,37,38,39,40,41,42,43,44,45,46] suffer from one or more of the following disadvantages: (i) inability to realize various filtering responses in all four possible modes; (ii) use of a greater number of active components; (iii) use of an excessive number of passive components; (iv) use of ungrounded passive elements; (v) need of some external switches; (vi) lack of built-in tuning capability; (vii) inability to control ω_o and Q independently; (viii) use of a complex active building block; (ix) need for inverting-type or double-type input signals.

Due to its simple structure, versatility, and CMOS integrability, the voltage differencing buffered amplifier (VDBA) is an alternative and suitable active building block for biquad filter solutions [47]. Interestingly, the internal circuit architecture of the VDBA block consists of an operational transconductance amplifier (OTA) and a voltage follower (VF) [48,49]. This simple circuitry implementation leads to low power consumption and small chip area requirements. Therefore, in this work we adopt the advantages provided by the VDBA device to design a mixed-mode universal biquad filter. The designed filter topology possesses the following salient properties: (i) use of a reasonable number of active and passive elements (i.e., two VDBAs, two resistors, and two capacitors); (ii) capability of realizing universal biquadratic filter functions in all four modes; (iii) employment of all grounded passive elements, except for VM; (iv) exhibits inbuilt tuning capability; (v) noninteractive control of Q; (vi) low-output impedance for VM and TIM operations. The functionality of the circuit has been evaluated through simulation results based upon TSMC 0.18-µm 1P6M CMOS technology parameters, and furthermore through the experimental measurements of the commercially available integrated circuit (IC), LT1228. Additionally, all properties of the proposed mixed-mode filter are mentioned and compared with the previous related works in Table 1. Furthermore,

Table 2. Performance comparison of the proposed filter with the recently proposed VDBA-based biquad filters.

Related Works/ Year	Configuration	Number of Components Used		Filter Functions Realized				Grounded Passive Elements	Inbuilt Tunability	Independent Control of ωo and Q	Need for Inverting or Double Input Signal(s)
		Active	Passive	VM	CM	TAM	TIM
[50]/2009	SIMO	FB-VDBA = 2	R = 4, C = 2	LP, BP, HP	--	BP, HP	--	no	yes	no	no
[51]/2012	MISO	VDBA = 2	Figure 3: C = 2	all five	--	--	--	no	yes	no	yes
			Figure 4: R = 1, C = 2	all five	--	--	--	no	yes	yes	no
[52]/2016	MISO	VDBA = 2	C = 2	all five	--	--	--	no	yes	no	yes
[53]/2016	MISO	VDBA = 2	C = 2	all five	--	--	--	no	yes	no	yes
[54]/2017	SISO	VDBA = 1	R = 3-4, C = 2	LP, BP, HP	--	--	--	no	yes	yes	no
[55]/2017	MIMO	VDBA = 2	C = 2	LP, BP, HP, BS	--	--	--	no	yes	no	no
[56]/2018	SIMO	DO-VDBA = 1	R = 2, C = 2	--	all five	--	--	no	yes	yes	no
[57]/2020	MISO	VDBA = 2	C = 2	all five	--	--	--	no	yes	yes	yes
[58]/2021	MISO	VDBA = 2	C = 2	LP, BP, HP, BS	--	--	--	no	yes	yes	no
Proposed circuit	MISO/ SIMO	VDBA = 2	R = 2, C = 2	all five	all five	all five	LP, BP	yes (except for VM)	yes	yes	no

Notes: FB-VDBA: fully balanced voltage differencing buffered amplifier, DO-VDBA: dual-output voltage differencing buffered amplifier.

presents a comprehensive comparison illustrating the superiority of the proposed mixed-mode universal filter over the earlier reported relevant VDBA-based biquad configurations [50,51,52,53,54,55,56,57,58]. As can be observed, no earlier VDBA-based filter realization can be operated in all four modes of operation. The passive components used for their realizations are all floating. Although the works proposed in [54,56] use a single VDBA as an active element, they suffer from operating in only a single mode and using at least four floating passive components.

The paper is organized as follows, Section 2 describes the VDBA. The proposed mixed-mode universal filter is proposed in Section 3. The non-ideal gain effect, sensitivity performance, and parasitic impedance effect are investigated in Section 4 and Section 5, respectively. The simulation results are given in Section 6, while the practical circuit implementation and the experimental results are presented in Section 7. Finally, the paper is concluded in Section 8.

2. VDBA Description

The electrical symbol of the VDBA is shown in Figure 1. The defining characteristic of the VDBA can be described by the following matrix equation:

$$\left[\begin{array}{c}{i}_p\\ i_n\\ i_z\\ v_w\end{array}\right]=\left[\begin{array}{cccc}0& 0& 0& 0\\ 0& 0& 0& 0\\ \alpha g_m& -\alpha g_m& 0& 0\\ 0& 0& \beta & 0\end{array}\right]·\left[\begin{array}{c}{v}_p\\ v_n\\ v_z\\ i_w\end{array}\right],$$

(1)

where g_m is the transconductance gain of the VDBA. The transconductance g_m, as usual, can be tuned by a bias current or voltage, thereby imparting tunability to the structure. Further, α and β are the non-ideal transconductance gain and nonideal voltage gain, respectively. These non-ideal gains can be defined as α = (1 + ε_α) and β = (1 + ε_β), in which the tracking errors are identified as |ε_α| << 1 and |ε_β| << 1. Accordingly, the values of α and β are ideally equal to unity.

As mentioned above, the VDBA block comprises two essential circuit blocks: an OTA and a VF [47,48]. The simple CMOS implementation of the VDBA used in this work is shown in Figure 2, in which the OTA consists of transistors M₁-M₆; and it is followed by a VF formed by transistors M₇–M₁₄. A pair of diode-connected PMOS active load (M₃–M₄) is driven by a source couple pair (M₁–M₂). The transconductance gain (g_m) of the OTA stage can be externally tuned by the bias current (I_B), as described by the following expression:

$$g_m=\sqrt{K_n\left(\frac{W}{L}\right)I_B},$$

(2)

where K_n = μ_nC_ox is the transconductance parameter, and (W/L) is the ratio of the width-to-length of the transistors M₁ and M₂. Note from Equation (2) that the transconductance g_m is electronically adjustable utilizing I_B.

Further, the voltage drop across the grounded impedance at terminal z (v_z) is then conveyed to the w terminal with a unity voltage gain by the VF. Thus, the negative-feedback loop established by M₇-M₁₁ provides a very low output impedance at the w terminal. For the simulation purpose, the TSMC 0.18-µm level 7 CMOS model parameter has been employed, where the transistor aspect ratios are given in

Table 3. Transistors’ aspect ratios in Figure 2.

Transistors	W(µm)/L(µm)
M1-M2, M5, M7-M8, M12-M13	2.4/0.18
M3, M9, M14	5/0.18
M4, M10	5.2/0.18
M6	3.25/0.18
M11	10/0.18

.

3. Proposed Mixed-Mode Universal Biquad Filter

The proposed configuration, which is realized by two VDBAs, two resistors, and two capacitors, is shown in Figure 3. It is important to note that, in this realization, the resistors R₁ and R₂ are permanently grounded. From the proposed circuit in Figure 3, the universal biquadratic filter operated in all four possible modes is available as follows.

⮚

For VM operation: Assuming ideal VDBA (i.e., α =β = 1) and setting i_in = 0, the general voltage biquadratic transfer functions of this MISO filter can be obtained as follows.

• With v_in = v₁ (input voltage) and v₂ = v₃ = v₄ = 0 (grounded), then the LP response is realized as:

  $$T_{LP(VM)}=\frac{v_{out}}{v_{in}}=\frac{\left(\frac{g_{m1}{g}_{m2}}{C_1{C}_2}\right)}{D(s)}.$$

  (3)
• With v_in = v₂, v₁ = v₃ = v₄ = 0, and g_m2 = 1/R₂, then the BP response is realized as:

  $$T_{BP(VM)}=\frac{v_{out}}{v_{in}}=\frac{\left(\frac{g_{m2}}{C_2}\right)s}{D(s)}.$$

  (4)
• With v_in = v₄, and v₁ = v₂ = v₃ = 0, then the HP response is realized as:

  $$T_{HP\left(VM\right)}=\frac{v_{out}}{v_{in}}=\frac{s^2}{D\left(s\right)}.$$

  (5)
• With v_in = v₁ = v₄, and v₂ = v₃ = 0, then the BS response is realized as:

  $$T_{BS\left(VM\right)}=\frac{v_{out}}{v_{in}}=\frac{s^2+\left(\frac{g_{m1}{g}_{m2}}{C_1{C}_2}\right)}{D\left(s\right)}.$$

  (6)
• With v_in = v₁ = v₃ = v₄, v₂ = 0, and g_m2 = 1/R₂, then the AP response is realized as:

  $$T_{AP\left(VM\right)}=\frac{v_{out}}{v_{in}}=\frac{s^2-\left(\frac{g_{m2}}{C_2}\right)s+\left(\frac{g_{m1}{g}_{m2}}{C_1{C}_2}\right)}{D\left(s\right)}.$$

  (7)

  where

  $$D(s)=s^2+\left(\frac{s}{R_2{C}_2}\right)+\left(\frac{g_{m1}{g}_{m2}}{C_1{C}_2}\right).$$

  (8)
  Under appropriate conditions, the proposed circuit realizes all five generic biquadratic filter responses at v_out, which are taken from the w-terminal of VDBA2. Thus, the voltage output of the circuit has a very low output impedance, which is suitable for VM cascadability. Moreover, in this MISO configuration, there is no requirement for negative and double input voltage signals to realize the desired filter responses.

⮚

For CM operation: If v₁ = v₂ = v₃ = v₄ = 0 (grounded), the CM biquad transfer functions for this SIMO filter, attained from the circuit analysis of Figure 3, are given by

$$T_{LP\left(CM\right)}=\frac{i_{LP}}{i_{in}}=\frac{-H_0\left(\frac{g_{m1}{g}_{m2}}{C_1{C}_2}\right)}{D\left(s\right)},$$

(9)

$$T_{BP\left(CM\right)}=\frac{i_{BP}}{i_{in}}=\frac{\left(\frac{s}{R_2{C}_2}\right)}{D\left(s\right)},$$

(10)

and

$$T_{HP\left(CM\right)}=\frac{i_{HP}}{i_{\mathrm{in}}}=\frac{s^2}{D\left(s\right)},$$

(11)

where H₀ is the passband gain equal to 1/g_m2R₁. Additionally, for R₁ = 1/g_m2, the BS current response can be realized by connecting the appropriate output currents as i_BS = i_HP – i_LP. In the same way, the AP response can also be obtained by the interconnection of LP, BP, and HP responses as i_AP = i_HP – i_BP – i_LP.

⮚

For TAM operation: With v_in = v₃ and v₁ = v₂ = v₄ = 0, then we obtain the TAM filter functions as follows:

$$T_{\mathit{LP}\left(\mathit{TAM}\right)}=\frac{i_{\mathit{LP}}}{v_{\mathit{in}}}=\frac{H_1\left(\frac{g_{m1}{g}_{m2}}{C_1{C}_2}\right)}{D\left(s\right)},$$

(12)

$$T_{\mathit{BP}\left(\mathit{TAM}\right)}=\frac{i_{\mathit{BP}}}{v_{\mathit{in}}}=\frac{-H_2\left(\frac{s}{R_2{C}_2}\right)}{D\left(s\right)},$$

(13)

$$T_{\mathit{HP}\left(\mathit{TAM}\right)}=\frac{i_{\mathit{HP}}}{v_{\mathit{in}}}=\frac{-H_2{s}^2}{D\left(s\right)},$$

(14)

$$T_{\mathit{BS}\left(\mathit{TAM}\right)}=\frac{\left(i_{\mathit{LP}}-i_{\mathit{HP}}\right)}{v_{\mathit{in}}}=\frac{H_2\left(s^2+\frac{g_{m1}}{R_1{C}_1{C}_2}\right)}{D\left(s\right)},$$

(15)

and

$$T_{\mathit{AP}\left(\mathit{TAM}\right)}=\frac{\left(i_{\mathit{LP}}+i_{\mathit{BP}}-i_{\mathit{HP}}\right)}{v_{\mathit{in}}}=\frac{H_2\left(s^2-\frac{s}{R_2{C}_2}+\frac{g_{m1}}{R_1{C}_1{C}_2}\right)}{D\left(s\right)}.$$

(16)

Equations (12)–(16) represent the TAM filter functions of the LP, BP, HP, BS, and AP responses with controllable passband gains, respectively. Gain constants can be defined as H₁ = 1/R₁ and H₂ = g_m2. It should also be noted from Equations (15) and (16) that a simple component matching condition (R₁ = 1/g_m2) is required in the case of BS and AP filter realizations.

⮚

For TIM operation: With all input voltages kept grounded (v₁ = v₂ = v₃ = v₄ = 0), the configuration in Figure 3 now works in TIM. For this operation, the circuit will realize only two LP and BP biquad filter functions without the requirement of any component matching constraints. The TIM transfer functions related to the outputs v_out and v_o(TIM) of the circuit are given by

$$T_{\mathit{LP}\left(TIM\right)}=\frac{v_{o(TIM)}}{i_{\mathit{in}}}=\frac{-\left(\frac{1}{H_2}\right)\left(\frac{g_{m1}{g}_{m2}}{C_1{C}_2}\right)}{D\left(s\right)},$$

(17)

and

$$T_{\mathit{BP}\left(TIM\right)}=\frac{v_{\mathrm{out}}}{i_{\mathit{in}}}=\frac{H_3\left(\frac{s}{R_2{C}_2}\right)}{D\left(s\right)},$$

(18)

where H₃ = R₂.

In all the above working modes, the important filter characteristics ω_o and Q according to Equation (8) are found as:

$${\omega }_o=2\pi f_o=\sqrt{\frac{g_{m1}{g}_{m2}}{C_1{C}_2}},$$

(19)

and

$$Q=R_2\sqrt{\frac{g_{m1}{g}_{m2}{C}_2}{C_1}}.$$

(20)

Inspection of Equations (19) and (20) reveals that the characteristic frequency ω_o can be tuned electronically through the transconductance g_mi (i = 1, 2) of the corresponding VDBA. Moreover, the filter parameter Q is independently controllable by the R₂. Hence, the high-Q filter could be conveniently obtained by simply adjusting a single resistance R₂.

4. Analysis of the Non-Ideal Gain Effect and Sensitivity Performance

Considering only the influence of the non-ideal gains (α =β ≠ 1), the characteristics ω_o and Q of the proposed filter will be modified as:

$${\omega }_o=\sqrt{\frac{{\alpha }_1{\alpha }_2{\beta }_1{g}_{m1}{g}_{m2}}{C_1{C}_2}},$$

(21)

and

$$Q=R_2\sqrt{\frac{{\alpha }_1{\alpha }_2{\beta }_1{g}_{m1}{g}_{m2}{C}_2}{C_1}},$$

(22)

where α_i and β_i (i = 1, 2) are the parameters α and β of the i-th VDBA, respectively.

The sensitivity analysis of ω_o and Q with respect to active and passive components is also carried out, and the calculation results are obtained as:

$$S_{{\alpha }_1}^{{\omega }_o}=S_{{\alpha }_2}^{{\omega }_o}=S_{{\beta }_1}^{{\omega }_o}=S_{g_{m1}}^{{\omega }_o}=S_{g_{m2}}^{{\omega }_o}=\frac{1}{2},$$

(23)

$$S_{C_1}^{{\omega }_o}=S_{C_2}^{{\omega }_o}=-\frac{1}{2},$$

(24)

$$S_{{\alpha }_1}^Q=S_{{\alpha }_2}^Q=S_{{\beta }_1}^Q=S_{g_{m1}}^Q=S_{g_{m2}}^Q=\frac{1}{2},$$

(25)

and

$$S_{R_2}^Q=1\begin{array}{c}\end{array},\begin{array}{c}\end{array}{S}_{C_1}^Q=-S_{C_2}^Q=-\frac{1}{2}.$$

(26)

It can be easily deduced that all the sensitivity coefficients of ω_o and Q are not greater than one in all four modes of operation.

5. Analysis of the Parasitic Impedance Effect

In this section, the effect of various parasitic impedances of the employed VDBA on the performance of the proposed mixed-mode universal filter in Figure 3 is to be analyzed. In practice, the non-ideal VDBA model with its various terminal parasitics is represented in Figure 4. It appears that the finite parasitic resistances and capacitances at the p, n, and z terminals are in the form [R_p//(1/sC_p)], [R_n//(1/sC_n)], and [R_z//(1/sC_z)], respectively, while the low-value serial resistance (R_w) appears at the w terminal. Ideally, these parasitic values are assumed to be R_p = R_n = R_z = ∞, R_w = 0, and C_p = C_n = C_z = 0. Under the effect of these parasitics, the non-ideal denominator of all transfer functions in all four working modes becomes:

$$D_n(s)=\left(s^2{ R\prime }_2{R}_{z1}{ C\prime }_1{ C\prime }_2+s{R}_{z1}{ C\prime }_1+s{ R\prime }_2{ C\prime }_2+1\right)\left(s{R}_{w1}{C}_{p2}+1\right)+g_{m1}{g}_{m2}{ R \prime }_2{R}_{z1},$$

(27)

where R′₂ = R₂ // R_z2 // R_n1, C′₁ = C₁ + C_z1, and C′₂ = C₂ + C_z2 + C_n1. Equation (27) illustrates that the order of the filter function is modified due to the parasitic pole ω_parasite, (i.e., ω_parasite = 1/R_w1C_p2). However, this effect can be diminished if the proposed circuit is designed to operate at a useful frequency much less than ω_parasite or under the following condition: ω << 0.1 ω_parasite. As the term (sR_w1C_p2 + 1) is made close to unity, Equation (27) can be further simplified to

$$D_n(s)\cong s^2+\left(\frac{1}{{ R\prime }_2{ C\prime }_2}+\frac{1}{R_{z1}{ C\prime }_1}\right)s+\left(\frac{g_{m1}{g}_{m2}+\frac{1}{{ R \prime }_2{R}_{z1}}}{{ C\prime }_1{ C\prime }_2}\right).$$

(28)

From D_n(s), the expressions for ω_o and Q in the presence of parasitic impedances are thus obtained as:

$${\omega }_o=\sqrt{\frac{g_{m1}{g}_{m2}+\frac{1}{{ R \prime }_2{R}_{z1}}}{{ C\prime }_1{ C\prime }_2}},$$

(29)

and

$$Q=\left(\frac{{ R\prime }_2{R}_{z1}{ C\prime }_1}{R_{z1}{ C\prime }_1+{ R\prime }_2{ C\prime }_2}\right)\sqrt{\frac{\left(g_{m1}{g}_{m2}+\frac{1}{{ R \prime }_2{R}_{z1}}\right){ C\prime }_2}{{ C\prime }_1}}.$$

(30)

Therefore, it may be concluded that the parasitic effects on the ω_o and Q would be alleviated if the following designs must be satisfied:

maximum (R₁, R₂) << parasitic resistances (R_n1, R_p2, R_z2),

(31)

and

minimum (C₁, C₂) >> parasitic capacitances (C_n1, C_z1, C_z2).

(32)

6. Simulation Results

The functionality of the proposed mixed-mode universal filter in Figure 3 was validated by the PSPICE circuit simulation program. The VDBA was modeled using the CMOS structure mentioned in Figure 2 with ±V = 0.75 V and I_A = 15 µA. In all simulations, the capacitor values were chosen with C₁ = C₂ = 50 pF. The circuit was designed for f_o = ω_o/2π = 1.52 MHz and Q = 1; the active and passive components were chosen as: g_m1 = g_m2 = 0.48 mA/V (I_B1 = I_B2 = 50 µA), and R₁ = R₂ = 2 kΩ. Figure 5 and Figure 6 illustrate the ideal and simulated LP, BP, HP, BS, and AP frequency responses for VM and TAM (i.e., when the input is voltage), respectively. Figure 7 shows the ideal and simulated LP, BP, and HP gain responses for CM and LP and BP in TIM (i.e., when the input is current). The simulated f_o of the BP filter was measured as 1.44 MHz, which is an error of 5.26% concerning its theoretical value. The simulation results of Figure 6 also show that the passband gain H₁ of the LP response for TAM is obtained as −66 dBS, which depends on H₁ = 20 log₁₀ (1/R₁). Similarly, the passband gains H₂ for BP, HP, BS, and AP responses are the same as the gain H₁ of the LP filter because of H₂ = 20 log₁₀ (g_m2) due to g_m2 = 1/R₁.

To examine the transient behavior of the proposed filter, the LP, BP, and HP responses were carried out for the VM operation. The sinusoidal input voltage of 50 mV (peak) at a frequency of 1.52 MHz was applied and the corresponding output current waveforms are given in Figure 8. As can be monitored, the phase differences between the input and LP, BP, and HP outputs are found to be −92.73°, 5.45°, and 87.29°, which are consistent with ideal values equal to −90° 0°, and 90°, respectively. The percentages of the total harmonic distortion (THD) for the three filter outputs are 0.22% for LP, 1.12% for BP, and 0.64% for HP. In addition, the THD variations of the LP, BP, and HP output voltages on the input signal amplitudes are also shown in Figure 9. It is shown that when the applied input signal amplitude increases by 100 mV (peak), the THD values are within 2.2%. Through the simulation results, the circuit has a total power consumption of 0.373 mW.

As indicated in Equations (19) and (20), the parameters ω_o and Q of the proposed filter can be set orthogonally. Figure 10 shows the Q-factor adjustability of the BP responses in VM for various values of R₂. In this case, the Q-factors are set as 0.5, 2.4, 9.5, and 95.5 with the R₂ value of 1 kΩ, 5 kΩ, 20 kΩ, and 200 kΩ, respectively. The results demonstrate that the high-Q tuning can be achieved by adjusting R₂ without influencing f_o. Figure 11 represents the VM gain responses of the BP filter for three different values of I_B and R₂. The BP filter is designed for f_o = 1.12 MHz, 2.15 MHz, and 3.72 MHz, while keeping Q fixed at 9.5.

Table 4. Details of component settings used to obtain a specified f_o in Figure 11.

IB = IB1 = IB2 (µA)	gm = gm1 = gm2 (mA/V)	R2 (kΩ)	fo (MHz)		Deviation in fo (%)
			Ideal Value	Simulated Value
30	0.37	25.7	1.12	1.09	2.67
100	0.67	14	2.15	2.24	4.18
300	1.17	8.12	3.72	3.52	5.38

gives the component values used in Figure 11 and the corresponding calculated and simulated f_o.

To study the effect of temperature variations, the proposed filter was analyzed under various ambient temperatures. Figure 12 demonstrates the simulated frequency responses of the AP filter in VM for different temperatures (0 °C, 20 °C, 50 °C, 75 °C, and 100 °C). At the natural angular frequency f_o = 1.52 MHz, the simulation results show that the gain and phase responses lie within the range of –1.3 dBV to –2.7 dBV, and –184° to –228°, respectively. This variation does not have a strong effect on the gain and phase responses of the circuit. The noise behavior of the proposed filter versus the frequency has also been evaluated, as shown in Figure 13. The output voltage noises of the BP filter at the frequency of 1.52 MHz were found to be 20.50 nV/Hz^1/2 for VM and TIM operations, while the output current noises for CM and TAM were 8.45 pA/Hz^1/2.

The Monte Carlo statistical analysis of the proposed filter is next performed to perceive the effects of the passive component deviations on the filter performance. Statistical analysis with 5% random deviation in both resistor and capacitor values was performed simultaneously for 200 samples. The results for LP, BP, and HP responses in VM operation are achieved as in Figure 14. Additionally, the corresponding histogram demonstrating the f_o variations in BP output is shown in Figure 15. According to the statistical results, the mean, median, and standard deviation were, respectively 1.50134 MHz, 1.49936 MHz, and 53.2151 kHz, which implies that the proposed filter exhibits a reasonable sensitivity figure to the passive component tolerances. This further validates the robustness of the design.

7. Experimental Results

The features of the proposed mixed-mode universal filter configuration in Figure 3 were also verified by laboratory experiments using a commercially available IC LT1228 from Linear Technology [59]. Figure 16 shows the PCB realized for measurement purposes. The supply voltage used was ±5 V. The experimental setup of the proposed mixed-mode universal filter utilizing the PCB board in Figure 16 is also shown in Figure 17. In CM and TIM measurements, an additional AD844 and a conversion resistor R_C were employed to perform the voltage-to-current conversion (V-to-I), where R_C = 1 kΩ. On the other hand, to obtain CM and TAM filter results, two AD844s and a resistor R_C were employed as a current-to-voltage converter (I-to-V). The passive and active components were selected as R₁ = R₂ = 1 kΩ, C₁ = C₂ = 100 pF, and g_m1 = g_m2 = 1 mA/V (I_B1 = I_B2 = 100 µA, where g_mi = 10 I_Bi). As a consequence, the theoretical filter parameters for this design were f_o = 1.59 MHz and Q = 1. Figure 18 shows the experimental measurements in the time domain of the input and output responses in VM operation, for a 50 mV (peak) sinusoidal input voltage (v_in) at 1.59 MHz. The corresponding spectral analyses of the v_out were also measured, and the results are provided in Figure 19. The measured results indicate that the THD figures for the LP, BP, HP, BS, and AP output responses were found to be 1.23%, 2.05%, 1.78%, 0.87%, and 2.04%, respectively. Hence, they have no significant distortion that can be observed in our frequency range of interest. The experimental results of Figure 19 also show that the spurious-free dynamic range (SFDR) for the cases of LP, BP, HP, BS, and AP were determined to be 40.70 dBc, 34.60 dBc, 38.07 dBc, 44.82 dBc, and 34.66 dBc, respectively.

Furthermore, the ideal and experimental results of the frequency-domain responses obtained from the VM, CM, TAM, and TIM filters are given in Figure 20, Figure 21, Figure 22 and Figure 23, respectively. The results of Figure 20, Figure 21, Figure 22 and Figure 23 show that a good agreement between experimental measurements and theoretical predictions can be observed, as desired. Additionally, the experimental THD variations of the BP output in all modes of operation are plotted for various input signal amplitudes at f = 1.59 MHz, as given in Figure 24.

8. Conclusions

In this work, a mixed-mode universal filter configuration has been proposed based on only two VDBAs, two grounded resistors, and two capacitors. The proposed circuit is capable of realizing all five biquadratic filtering functions in VM, CM, and TAM operation. In TIM operation, the circuit can realize LP and BP responses. The circuit satisfies the major advantages simultaneously such as (i) employment of grounded passive components, except for VM operation; (ii) having electronic tunability for ω_o; (iii) independent controllability of its quality factor; (iv) unemploying inverting-type or double-type input signals; (v) having low output impedance for VM and TIM operations; (vi) low active and passive sensitivity features. The high-Q filter can be easily achieved through a single resistance adjustment. The mathematical analyses such as non-ideal gains, sensitivity performance and parasitic analysis along with the numerical simulation results and experimental measurement results are shown, in order to strengthen the design idea.